Damage Assessment of a Full-Scale Six-Story
Wood-Frame Building Following Triaxial
Shake Table Tests
John W. van de Lindt, M.ASCE1; Rakesh Gupta, M.ASCE2; Shiling Pei, M.ASCE3;
Kazuki Tachibana4; Yasuhiro Araki5; Douglas Rammer, M.ASCE6; and Hiroshi Isoda7
Abstract: In the summer of 2009, a full-scale midrise wood-frame building was tested under a series of simulated earthquakes on the world’s
largest shake table in Miki City, Japan. The objective of this series of tests was to validate a performance-based seismic design approach by
qualitatively and quantitatively examining the building’s seismic performance in terms of response kinematics and observed damage. This
paper presents the results of detailed damage inspections following each test in a series of five shake table tests, and explains their qualitative
synthesis to provide design method validation. The seismic test program had two phases. Phase I was the testing of a seven-story mixed-use
building with the first story consisting of a steel special moment frame (SMF) and stories 2–7 made of light-frame wood.
In Phase II, the SMF was heavily braced such that it effectively became an extension of the shake table and testing was conducted on only
stories 2–7, making the building a six-story light-frame multifamily residential building instead of a mixed-use building. All earthquake
motions were scalings of the 1994 Northridge earthquake at the Canoga Park recording station with seismic intensities ranging from peak
ground accelerations of 0.22 to 0.88 g. The building performed quite well during all earthquakes with damage only to the gypsum wall board
(drywall), no sill plate splitting, no nails withdrawing or pulling through the sheathing, no edge tearing of the sheathing, no visible stud
splitting around tie-down rods, and reasonable floor accelerations. On the basis of damage inspection, it was concluded that it is possible
to design this type of building and keep the damage to a manageable level during major earthquakes by utilizing the new design approach.
DOI: 10.1061/(ASCE)CF.1943-5509.0000202. © 2012 American Society of Civil Engineers.
CE Database subject headings: Damage; Earthquakes; Shake table tests; Full-scale tests; Experimentation; Multi-story buildings; Wood
structures.
Author keywords: Damage assessment; Earthquake; Shake table; Full-scale experiment; Performance.
Introduction
It is estimated that 80–90% of all structures in the United States are
wood structures (Malik 1995). In California, virtually all singlefamily dwellings are wood-frame construction and in Los Angeles
County, 96% of all buildings are wood-frame construction [Consortium of Universities for Research in Earthquake Engineering
(CUREE) 1998]. Wood-frame construction is not only used for single- and multifamily dwellings, but also for low-rise commercial
and industrial buildings. Historically, wood structures have performed extremely well with regard to protecting their occupants’
1
Professor and Garry Neil Drummond Endowed Chair, Dept. of Civil,
Construction, and Environmental Engineering, Univ. of Alabama, Tuscaloosa, AL (corresponding author). E-mail: jwvandelindt@eng.ua.edu
2
Professor, Dept. of Wood Science and Engineering, Oregon State
Univ., Corvallis, OR.
3
Assistant Professor, Dept. of Civil and Environmental Engineering,
South Dakota State Univ., Brookings, SD.
4
Ph.D. Candidate, Univ. of Tokyo, Tokyo, Japan.
5
Professor, Kobe Univ., Kobe, Japan.
6
Research Engineer, U.S. Forest Products Laboratory, Madison, WI.
7
Associate Professor, Shinshu Univ., Nagano, Japan.
Note. This manuscript was submitted on August 10, 2010; approved on
December 27, 2010; published online on December 30, 2010. Discussion
period open until July 1, 2012; separate discussions must be submitted for
individual papers. This paper is part of the Journal of Performance of
Constructed Facilities, Vol. 26, No. 1, February 1, 2012. ©ASCE, ISSN
0887-3828/2012/1-17–25/$25.00.
safety during seismic events because of their high strength to
weight ratio and highly nonlinear ductile behavior during
earthquakes that enables them to dissipate energy. However, the
energy-dissipating nonlinear behavior at times results in a level of
damage that society deems unacceptable, i.e., the 1994 Northridge
earthquake resulted in approximately US$40 billion in damage
with half of that amount to wood-frame buildings, though most
of this damage was in the nonstructural gypsum wallboard (GWB)
(Schierle 2002a, b).
NEESWood was a four-year, five-university project that sought
to develop a new design approach for taller wood-frame buildings
in earthquake-prone areas. The project started in 2005 with the
benchmark test of a full-scale two-story wood-frame townhouse
on two triaxial shake tables acting in unison at the University of
Buffalo Network for Earthquake Engineering Simulation (NEES)
site (Christovasilis et al. 2007). The goal of the benchmark testing
program was focused on the various construction elements that may
have influenced the seismic response of wood-frame buildings and
that should be considered in a performance-based seismic design.
Several seismic tests were conducted at different stages of construction to examine this issue. The GWB was repaired between
tests but sill plates were not repaired. Visual damage inspection
was conducted after each seismic test and observations were reported in Christovasilis et al. (2007). Different damage states were
correlated with the peak interstory drift recorded near the damaged
location. For a low interstory drift (0.1–0.5%), hairline cracking
of the sill plate was observed. This cracking grew and led to significant splitting of the first-floor sill plates at higher levels of
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interstory drift (greater than 2%), as one might expect. At this level,
cracking was also observed in vertical studs connected to holddowns. The GWB damage primarily included diagonal cracking
at the corners in which there were wall openings, crushing of GWB
corners, and buckling of GWB. Significant cracking and spalling of
stucco was also observed all around the building. The most significant structural damage was the splitting of sill plates of the narrow
wall piers of the garage. Correlations between interstory drift and
observed damage in the 2006 benchmark building test were used as
the various targets in the new performance-based seismic design
(PBSD) approach, namely simplified direct displacement design
(DDD) (Pang et al. 2010).
With the structural damage correlated to interstory drift, damage
control in PBSD was believed to be achievable by limiting interstory drifts in midrise wood-frame building design. However, it was
felt that this belief might be conservative, because the correlation
between damage and interstory drift used in the design process was
from a two-story building and the test in Japan was conducted on a
much taller building. The method mentioned previously was developed by Pang and Rosowsky (2007) and built on the earlier studies
for displacement-based design; see e.g., Priestley (1998) and
Filiatrault and Folz (2002). Table 1 shows seismic intensities used
in the Capstone test program. The detailed structural design, including shear transfer details and (continuous anchor tie-down) system
design, was conducted after the DDD shear wall selection procedure using the Seismic Analysis Package for Wood-frame Structures (SAPWood) software (SAPWood for Windows Version 1.0).
Seismic Test 2 had a hazard of 7% probability of exceedance in
50 years (7%=50) in an effort to engage the steel special moment
frame to a greater extent than the 10%=50 was able to achieve in
pretest computer simulations.
This paper presents the results of damage inspections following
each test in a series of five shake table tests and explains their qualitative synthesis to provide design method validation for the DDD
procedure. Damage is described qualitatively whereas response
kinematics are described quantitatively. For each seismic intensity
level shown in Table 1, a conclusion was reached as to whether the
performance was better than expected, as expected, or poorer than
expected.
Brief Description of Test Specimen
The Capstone test building was a six-story wood-frame apartment
building with one additional steel moment frame (SMF) story at the
bottom and a floor plan representative of a typical multistory residential condominium in California. It was constructed at full size
with 23 living units for the wood portion providing approximately
1;340 m2 (14;400 ft2 ) of residential living space. The bottom story
SMF had 223 m2 (2;400 ft2 ) of commercial retail space. Added
mass consisted of 64 two-ton steel plates that were used to bring
the test building to the design weight, which included dead load and
applicable live loads. The dead load was estimated on the basis of a
force-based design of the same architectural plan according to the
International Building Code [International Code Council (ICC)
2009], including finishing materials such as floor tiles, insulation,
air conditioning units, wiring, and plumbing. The total weight of
the wood-only six-story building was 285 metric tons (628 kips).
The total weight of the seven-story wood-steel hybrid building was
361 metric tons (797 kips). The test building was standard lightframe construction with several notable exceptions: (1) the stud
packs were significantly larger than typical because of the height
of the building and the seismic intensity used in the design, and
(2) glulams were used (as drag struts) for all wood shear walls
to transfer shear throughout the building. These glulams also served
as headers over openings when needed. The first story had a clear
height of 2.75 m (9 ft) and the other five stories had a clear height of
2.44 m (8 ft). Detailed information about the test building can be
found in the NEESWood report by Pei et al. (2010).
There was no exterior finish material installed on the building,
but an equivalent amount of mass was added to simulate the weight
of exterior vinyl siding. It was felt after discussion with the project
advisory committee that vinyl siding would not provide additional
stiffness or strength to the specimen and could be neglected. Testing with exterior stucco was conducted by Filiatrault et al. (2010)
and provided a significant increase in both strength and stiffness,
thereby improving the overall performance of the building at all
seismic test levels. For all interior walls, 13-mm (1=2 in:)-thick
GWB was installed according to the California Building Code
[California Building Standards Commission (CBSC) 2007] Table
25-G with #6 drywall screws at 300-mm (16-in.) spacing on both
sides (i.e., not a “float” drywall installation) except for walls in the
stairwell (which only had drywall on one side) and the double midply walls. The GWB has historically been considered a nonstructural element in wood-frame design. However, damage assessment
after the 1994 Northridge earthquake suggested that most of the
loss was because of cracking and tearing of the GWB. Nails pulling
out of the oriented strand board (OSB) also contributed to failures
(Schierle 2002a, b). The drywall panels were purchased in Japan
and were “normal” strength Japanese drywall panels (drywall in
Japan is available in three different strengths). The drywall was installed with tape and putty on all joints except the wall-to-ceiling
joints and corners. Finishing as many joints as possible was desirable to provide realistic damage inspection results. The elevation
views of the test building are shown in Fig. 1. To identify damage
to shear walls, each shear wall was provided an identifier, which is
shown in Fig. 2. Over 300 channels of instrumentation were used to
record the building response kinematics during each test. Fig. 3
shows an example of a diagonally mounted string potentiometer
which was positioned on many of the shear walls to record deformation diagonally across the sheathing panel as a result of shear.
The absolute displacements were measured using 50 optical
tracking lights combined with seven high-resolution cameras as
shown in Fig. 4. Thus, absolute displacement was only known
for points on the exterior of the building and, thus, interior walls
Table 1. Seismic Intensities Used in Capstone Test Program
PGA (g)
Seismic test
1
2
3
4
5
Test date
Structure
Hazard level (%)
Scaling factor
X
Y
Z
June 30, 2009
Hybrid
July 6, 2009
Wood only
50=50 years
7=50 years
50=50 years
10=50 years
2=50 years
0.53
1.40
0.53
1.20
1.80
0.19
0.50
0.19
0.43
0.65
0.22
0.58
0.22
0.50
0.75
0.26
0.69
0.26
0.59
0.88
July 14, 2009
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Fig. 1. Test building elevations
Fig. 2. Shear wall identification scheme
connected at an exterior wall line were assumed to approximately
follow that displacement.
Description of Test Program
Recall that the Capstone test program consisted of two phases with
five shakes in total, as presented in Table 1. The input ground motions were four scaled versions of the Canoga Park record from the
1994 Northridge earthquake, as shown in Fig. 5.
All five tests were triaxial tests that simulated all the ground
motion components. There were no repairs or modifications of
the structure during the entire testing program; therefore, any reported structural and or nonstructural damage includes propagation
from previous tests, i.e., cumulative damage reporting over the entire study. This was not possible with the shake table occupation
time provided for the project, because the building had a finished
area equivalent to 1,200 standard GWB panels.
Test Results
This study focused on damage to the building and thus, only drift
results are presented here. For other detailed response results, such
Fig. 3. Diagonal deformation measurements using stringpot
as forces and accelerations, the interested reader is referred to Pei
et al. (2010). Table 2 presents the peak interstory drifts for each
story, which was computed by averaging the seven optical tracking
displacement measurements at each story diaphragm. Each row
varies by story, and each column by seismic test for both horizontal
directions. Table 3 presents these individual point interstory drifts
that can be assumed to approximately represent the peak interstory
drift for a single shear wall near that point. Torsional response of
the building was observed to result in peak interstory drifts for individual walls (Table 3) significantly higher than the peak interstory
drifts for the entire story (Table 2). For example, the peak interstory
drift for the entire story for all tests and all story levels is 1.88%
(Story 6, Seismic Test 5 in Table 2), whereas the peak interstory
drift for an individual wall was 3.08% (Table 3) at the same location, thus indicating the presence of torsion in the building.
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Fig. 4. Optical tracking system to record absolute displacements during testing
Fig. 5. Acceleration response spectra of unscaled Canoga Park record
for 5% damping
Damage Inspection and General Observation
An inspection group of approximately 40 people performed damage inspection immediately following each test. Teams of two people were each assigned one quadrant of one story in the building.
Different colored felt-tip markers, similar to the marking schemes
used in typical concrete seismic testing, were used after each test to
show the propagation of GWB cracks as a result of subsequent
shakes. No edge tearout of GWB was primarily attributed to the
fact the all edges of GWB had large edge distances. These large
distances were possible because it was an engineered building
(as opposed to a prescriptively built wall, in which generally only
one stud is behind one or two edges of GWB; hence, small-edge
distances for fasteners) and each GWB edge had more than one
stud behind it providing large edge distances. Overall damage
was limited to what has historically been described as nonstructural
damage, i.e., cracks in GWB. Most of the cracking was found near
window and door openings and propagated diagonally outward,
similar to typical damage found in GWB following a moderate
earthquake (Schierle 2002a, b). Fig. 6 shows typical cracks
observed as a result of the five shakes. Sill plates did not split anywhere in the building, which is unusual for this ground motion
intensity level. This is believed to be the result of the 6-mm
(1=4 in:)-diameter self-tapping screws used to anchor the shear
wall sill plates through the floor sheathing and into glulams,
and served as shear collectors rather than the typical 16 mm
(5=8 in:) diameter bolts. Fig. 7(a) shows the end of the sill plates
for one wall on each story that experienced average or above average drift. The slight damage seen to the Story 3 sill plate was the
Table 2. Maximum Interstory Drift (%) for All Tests
Seismic test →
Direction → Story ↓
1
2
3
4
5
6
7
1
2
3
4
5
X
Y
X
Y
X
Y
X
Y
X
Y
0.19
0.35
0.41
0.35
0.36
0.33
0.38
0.32
0.38
0.58
0.41
0.45
0.35
0.29
0.34
0.60
0.77
0.75
0.92
0.83
0.96
0.51
0.91
1.14
1.20
1.31
1.15
0.65
0.12
0.26
0.35
0.29
0.30
0.36
0.40
0.10
0.44
0.42
0.54
0.44
0.46
0.21
0.16
0.49
0.63
0.64
0.77
0.64
0.88
0.28
0.77
1.05
1.02
1.22
1.14
0.58
0.31
0.84
0.97
0.89
1.10
1.00
1.35
0.34
1.12
1.46
1.64
1.48
1.88
1.11
Note: Values are average value at centroid of floor plan.
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Table 3. Maximum Interstory Drift (%) at Any Individual Wall Line for Each Story During Seismic Tests 1–5
Seismic test →
Direction → Story ↓
1
2
3
4
5
6
7
1
2
3
4
5
X
Y
X
Y
X
Y
X
Y
X
Y
0.43
1.70
1.88
0.66
0.73
0.94
0.82
0.45
1.37
2.04
0.78
0.77
0.63
0.65
0.70
1.48
1.87
1.28
1.40
1.43
1.40
0.69
1.11
1.50
1.63
1.64
1.98
0.90
0.56
0.91
1.25
0.69
0.71
0.82
0.78
0.37
0.64
0.82
0.83
0.76
0.80
0.63
0.58
1.09
1.20
1.21
1.69
1.29
1.18
0.40
1.02
1.41
1.52
1.69
1.90
0.83
0.97
1.40
1.90
1.57
1.62
1.82
1.78
0.52
1.50
2.10
2.08
2.35
3.08
2.18
Fig. 6. Example of cracking propagation from the corners of a window
opening after five simulated earthquake tests
result of toe-nailing during construction and was marked as pretest
damage. Fig. 7(b) shows the top of the wood screws after removing
OSB on one side of the shear wall following the final seismic test.
Other than the damage to GWB, no additional damage was observed, i.e., no nail withdrawal, no nail pull-through in the sheathing, and no visible stud splitting around tie-down rods. In a typical
shear wall, testing without GWB failures like these are seen. But
the full-scale, six-story Capstone building did not see any of these
failures. This is because in shear wall testing, shear deformation is
dominant, whereas in a full-scale and especially a six-story building, other deformations (such as bending and axial) are also
present. Also, tie-down rods that extended the whole height of
the building resisted most of the overturning forces.
Correlation of Observed Damage to
Intensity and Drift
Intensity Level Correlation
Although damage was limited to dry wall cracks only, correlation
of damage to the seismic intensity test level can be identified during
all five tests. In the test at Seismic Intensity Level 1, only very minor cracking was observed around the openings, as shown in Fig. 8.
In many of these cases, the cracks were small enough to have been
covered/filled with paint. As was anticipated, Seismic Intensity
Level 2þ, which slightly exceeded the design-basis earthquake
(DBE), caused more damage. The cracking was definitely detectable at many locations, but was still limited to the GWB. At this
seismic intensity level, it became apparent that the stories with the
larger interstory drift levels had longer, wider, and at times more
numerous GWB cracks. Fig. 9 shows one of the more noticeable
crack patterns that occurred above several doorways after Seismic
Test 2. The diagonal pen marking indicates a section of the GWB
that may have slightly pulled away, or in which the paper was loosened. Seismic Test 3 was a smaller shake, but with the steel SMF
locked down, i.e., testing only the six-story wood building. During
this small shake, many locations had no propagation of crack damage. For example, Fig. 10 shows a vertical crack above the doorway
that occurred during Seismic Test 2 but did not widen or spall during Seismic Test 3. Because of the way the tests were performed, it
is difficult to tell if the 50%=50-year earthquake used in Seismic
Test 3 would have caused any appreciable damage even to the
GWB. It is likely there would have been only hairline cracking such
as that shown in Fig. 11.
Seismic Test 4 (ST4) was a DBE level earthquake and resulted
in more GWB damage. The start of some GWB spalling can be
seen in the photograph. In general, Seismic Test 4 propagated
existing cracks and caused some smaller cracks to branch off from
the main cracks. Fig. 12 shows some new cracking near one of the
corner GWB screws, indicating significant racking in the panel
after ST4. The propagation discussed previously was observed routinely, as shown in Fig. 13. The “ST4” marking is for both the upward and downwardly propagating cracks. Repairs (structural or to
the GWB) between tests were not made; thus, conclusions and correlations discussed in this paper only seek to better understand the
trends.
The final test [Seismic Test 5 (ST5)] in the Capstone test program was a maximum credible earthquake (MCE) level corresponding to a 2%=50-year event, statistically giving a return
period of approximately 2,500 years. In ST5, crack propagation
from the top corner of an opening connected to another crack
propagation from a GWB screw. This was observed for walls that
experienced the largest interstory drifts, i.e., near 3%, but not all.
An example of this type of damage is shown in Fig. 14. In some
places a crushed corner was observed, as shown in Fig. 15. A more
interesting occurrence was the substantial cracks that were observed to be new and not propagating from existing cracks from
the previous tests. This only occurred as a result of ST5 and an
example is shown in Fig. 16.
Drift Correlation
An effort is made here to qualitatively correlate damage with drift.
Initially, Story 2 had a smaller interstory drift during each of the
tests than Story 6 (Tables 2 and 3), yet the amount of damage
was about the same at both stories. Figs. 17 and 18 show very typical damage for Story 2 after ST5. Fig. 17 shows some light spalling, but in general the cracks did not extend all the way to the panel
seam or nearby wall corners. Fig. 18 shows two cracks failing to
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Fig. 7. (a) Sill plates remaining intact (i.e., no splitting) following all five shakes; (b) close-up of sill plate after removing wall sheathing
Fig. 8. Minor crack on Wall E4, Story 2 (over window opening) after
Level 1 shaking
Fig. 9. Crack on Wall D1, Story 4 (over door opening) after Seismic
Test 2
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Fig. 10. No new crack on Wall 2A, Story 7 (over door opening) after
Seismic Test 3; the crack shown was developed during Seismic Test 2
Fig. 13. Crack on Wall 2A, Story 5 (over door opening) after Seismic
Test 4
Fig. 11. Crack on Wall A3, Story 2 (over window opening)
Fig. 14. Crack on Wall A3, Story 4 (over window opening) after Seismic Test 5
Fig. 12. New crack on Wall D1, Story 3 (corner crushing) after Seismic
Test 4
Fig. 15. Crack on Wall D2, Story 6 (corner crashing) after Seismic
Test 5
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Fig. 16. New crack on Wall 2A, Story 7 (over door opening) after
Seismic Test 5
Fig. 19. Story 6, Wall E1; cracks develop all the way through panel
after Seismic Test 5
Fig. 17. Wall E1; cracks did not extend all the way to the panel edge
after Seismic Test 5
Fig. 20. Story 6, Wall E2; cracks develop all the way through panel for
all corners after Seismic Test 5
Fig. 18. Story 2, Wall E2; cracks failing to connect together after Seismic Test 5
connect following ST5 at Story 2. For some of the damaged GWB
in this study, cracks tended to propagate until they connected to
another crack, particularly when there was significant interstory
drift caused by a combination of shear and bending. This was typical on lower stories of the building because the overall interstory
drifts were lower. Comparatively, consider Story 6 following the
series of five shakes. The cracks tended to propagate all the way
through the panel as shown in Fig. 19. Fig. 20 shows this from
a full-panel vantage point. Further, in Story 6, crushing of the panel
corners was more routinely observed, as shown in Fig. 21. Most of
the damage in lower stories was attributed to shear deformation,
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Fig. 21. Crushing of corners also seen at Story 6, Wall E5 after seismic
test
author(s) and do not necessarily reflect the views of the NSF.
The authors are grateful to the overall NEESWood project team
made up of David V. Rosowsky, Andre Filiatrault, Rachel A.
Davidson, and Michael D. Symans. Thank you also to Weichang
Pang of Clemson University for his participation in the design portion of the Capstone test specimen. Thank you to NSF EU’s Doug
Allen and Kathryn Pfretzschner; researchers Izumi Nakamura,
Chikahiro Minowa, and Professor Mikio Koshihara. Graduate student Tomoya Okazaki contributed to the construction and instrumentation. Thank you also to Steve Pryor and Tim Ellis of
Simpson Strong-Tie and David Clyne of Maui Homes USA. Technical collaborators beyond the authors’ affiliations included
FPInnovations Forintek Division and Maui Homes. Financial
and in-kind product and personal donations were provided by
Simpson Strong-Tie; Maui Homes; British Columbia Ministry of
Housing and Social Development; Stanley Bostitch; Strocal,
Inc.; Structural Solutions, Inc.; Louisiana-Pacific Corp.; Natural
Resources Canada; Forestry Innovation Investment; APA—The
Engineered Wood Association; the American Forest and Paper
Association; Howdy; Ainsworth; Calvert Glulam; and the 2 × 4
Association of Japan.
References
whereas in upper stories the damage was attributed to a combination of shear and bending.
Conclusions
This paper presents the results of damage inspections following
a series of simulated earthquake tests of a full-scale, six-story,
wood-frame building and qualitatively correlates the interstory drift
with damage. The building performed quite well during all earthquakes, including the MCE level earthquake corresponding to a
2%=50-year event with damage only to the nonstructural elements,
i.e., GWB (drywall). There was no damage to any wood components of the building, including no sill plate splitting, no nail withdrawal or nails pulling through the sheathing, no edge tearing of the
sheathing, and no crushing of the wood under tie-down rod-bearing
plates.
There was good correlation of the overall interstory drift with
damage. However, much of the drift in the upper building stories
was attributed to global bending of the building and not solely shear
deformation at the individual shear wall level. This results in a
blending (some portion shear and some portion bending) of drifts
between 1 and 3% as the story level increases in the building. However, there appears to be a general trend and thus correlating damage with overall interstory drift is an attainable goal, at least in the
less-than-3.5% interstory drift range, because a general correlation
was observed. Therefore, controlling drifts in engineering design
can work for damage control in midrise wood-frame buildings,
but should not be quantitatively extracted from shear wall tests
or low-rise shake table tests. The effect of preexisting damage
attributed to previous tests was neglected in the qualitative correlations discussed in this paper.
Acknowledgments
The material presented in this paper is based upon work supported
by the National Science Foundation (NSF) under Grant
No. CMMI-0529903 (NEES Research) and CMMI-0402490
(NEES Operations). Any opinions, findings, and conclusions or
recommendations expressed in this material are those of the
California Building Standards Commission (CBSC). (2007). California
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